Martensite and deformation twinning in austenitic steels

Materials Science and Engineering A273 – 275 (1999) 430 – 436
www.elsevier.com/locate/msea
Martensite and deformation twinning in austenitic steels
V. Tsakiris a, D.V. Edmonds b,*
a
Commercial and Logistics Department, Effem Argentina, 6608, Mercedes, Argentina
b
Department of Materials, Uni6ersity of Leeds, Leeds, LS2 9JT, UK
Abstract
The structural changes that occur in highly-alloyed austenitic steels during plastic deformation have been studied as a function
of temperature and plastic strain. Stress-assisted and strain-induced martensites can occur, but also, deformation twinning can be
identified by transmission electron microscopy. In the high-Mn austenite of Hadfield steel deformation is controlled by slip and
twinning over a wide temperature range. In high-Ni and more complex alloyed austenites (such as in TRIP steels) deformation
involves martensite formation, both stress-assisted and strain-induced, but near room temperature and above the influence of
mechanical twinning, is also apparent. © 1999 Elsevier Science S.A. All rights reserved.
Keywords: Austenitic steels; Plastic deformation; Martensite; Twinning
1. Introduction
Austenitic steels form an important group of industrial alloys with a broad range of properties. They
contain austenite stabilising elements, e.g. Mn or Ni
which open the g-field and at sufficient concentrations
preserve the fcc austenite phase at room temperature
and below. The response of this stable or metastable
austenite to deformation can result in enhanced properties, e.g. high work hardening or high tensile ductility,
useful in a range of industrial applications. However,
these properties are achieved by mechanisms involving
interaction between slip and, in the highly-alloyed
austenite, the potential for mechanical twinning, and
also, martensite transformation induced by the deformation. Consequently, the deformation microstructures
of these austenitic steels can be quite complex and the
problem for early metallographers was firstly to differentiate between mechanical twinning and martensite.
Mechanical twinning in fcc metals is less common but
can be assisted by a high solute concentration which
can simultaneously raise the shear stress for slip and
reduce the stacking fault energy. Thus deformation
* Corresponding author. Tel.: +44-113-233-2341; fax: +44-113233-2384.
E-mail address: [email protected] (D.V. Edmonds)
twinning has been reported to occur, for example, in
austenitic stainless steels [1–3].
Deformation twinning and deformation-induced
martensitic transformation differ in that the latter is
also driven by a chemical free energy change, but are
microstructurally similar in that both involve diffusionless shear of a constrained plate-shaped region of parent crystal which differentiates it from the surrounding
material. Additionally, they might not be expected to
have such dissimilar effects on the accompanying deformation behaviour and properties of the bulk alloy.
Early work on high-Mn Hadfield steel attributed a high
work-hardening rate to the formation of a- or omartensite but the consensus of later studies [4–9] was
that the microstructural striations observed were due to
deformation twinning, although it has been argued
more recently that the high work hardening is solely
due to dynamic strain ageing [10]. On the other hand,
the formation of martensite in high-Ni alloys or more
complex-alloyed austenitic steels is well documented
[11–17] although differentiation between strain-induced
martensite and bands of twins remains a difficulty
[14,15].
The present paper examines the deformation microstructures in three highly-alloyed austenites over a
wide test temperature and strain range, and compares
the observations and the mechanical behaviour.
0921-5093/99/$ - see front matter © 1999 Elsevier Science S.A. All rights reserved.
PII: S 0 9 2 1 - 5 0 9 3 ( 9 9 ) 0 0 3 2 2 - 6
V. Tsakiris, D.V. Edmonds / Materials Science and Engineering A273–275 (1999) 430–436
431
Table 1
Chemical compositions and approximate Ms and Md temperatures
Sample
Composition (wt.%)
Hadfield steel
High-Ni alloy
TRIP Steel
C
Si
Mn
Ni
Cr
Mo
0.96
0.6
0.29
0.78
–
2.02
12.85
–
0.81
–
22.8
7.7
–
–
8.9
–
–
4.09
2. Experimental procedures
Three steels were used, two of them based on Mn or
Ni alloying with the third more complex alloyed with
Ni, Cr, Mo and Si (the first composition simulates that
of a Hadfield steel and the last of a transformation
induced plasticity (TRIP) steel [16]). The steels were
manufactured as 20 kg vacuum melts, hot forged and
hot rolled to 10 mm diameter. Chemical analyses and
approximate Ms and Md temperatures are given in
Table 1. The samples were sealed in evacuated silica
capsules under a partial pressure of argon and heat
treated and water quenched according to Table 2 which
also gives the final grain sizes. Tensile specimens with a
17 mm gauge length and 3.5 mm gauge diameter were
tested in an Instron 1195 machine at a nominal strain
rate of 8.3×10 − 4 s − 1. Elevated temperature tests were
conducted using a temperature-controlled resistanceheated split-furnace with the specimen temperature
recorded directly by a thermocouple. Low temperature
tests employed immersion in liquid nitrogen (− 196°C),
a mixture of ethyl alcohol and dry ice (−25–
−74.5°C) and an ice – water mixture (0°C). Ms and Md
temperatures (Table 1) and the amount of martensite
formed were determined by measuring the saturation
magnetisation of tensile specimens before and after
tensile testing [18]. Specimens for light and transmission
electron microscopy were prepared according to customary practices by mechanical and electrolytic polishing and etching as detailed previously [18].
Ms (°C)
Md (°C)
B−196
−60
−196
B−196
100
35
strength and work hardening as a function of
temperature are presented in Fig. 1. The measure of
work hardening used is the difference in flow stress at
plastic strains of 0.04 and 0.002, and reflects the
particularly high work hardenening behaviour of this
steel in the range − 75– + 300°C. Fig. 2 shows the
temperature dependence of work hardening at a range
of plastic strain values and is equivalent to published
results over a smaller range of conditions [10] (Adler,
private communication, (1984).).
Fig. 3 shows the microstructure after 0.02 plastic
strain. Similar deformation microstructures have been
presented by others [4,10]. The long thin parallelsided deformation markings, consistent with (111) type
habit, variously described previously as stacking faults,
3. Results and discussion
For the high-Mn Hadfield steel the UTS, yield
Table 2
Heat treatments and final grain sizes
Sample
Heat treatment
Grain size (mm)
Hadfield steel
High-Ni alloy
TRIP Steel
1100°C for 30 min
1100°C for 60 min
1200°C for 60 min
170
100
280
Fig. 1. UTS, yield strength and work hardening as a function of
temperature for high-Mn austenite (Hadfield steel).
432
V. Tsakiris, D.V. Edmonds / Materials Science and Engineering A273–275 (1999) 430–436
Fig. 4. Electron micrograph of high-Mn austenite strained to fracture
at − 25°C.
Fig. 2. Temperature dependence of work hardening at different true
plastic strains for high-Mn austenite.
a- or o-martensite, or twins, increase with strain and
with decreasing temperature. Quantitative measurements indicated that these striations appear after a
critical strain (which increases with temperature) and
that their quantity increases parabolically and saturates
Fig. 3. Light micrograph of deformation microstructure in high-Mn
austenite strained 0.02 at room temperature.
after a certain plastic strain which decreases as the
temperature increases, similar to the kinetics of fcc
twinning [19]. Fig. 4 is a bright-field electron micrograph of the deformed structure and shows very thin
striations gathering into thicker bands along with a
high dislocation density. The analysis of Fig. 5 indicates
that the striations and alternate bands are twin related.
The beam direction used should identify o-martensite
reflections if present [9]. Magnetic measurements also
found the specimens to be fully austenitic after large
plastic strains to fracture. This behaviour is consistent
with measured Ms and Md temperatures below −
196°C. Consequently, the deformation markings are
confirmed to be (111) deformation twinning and not
martensite as occasionally reported in the past.
A maximum in work hardening around room temperature at low plastic strains is noticed in Fig. 2, which
has been attributed to a unique interaction between
dislocations and C–Mn couples to give dynamic strain
ageing [10], consistent with the serrated plastic flow
observed. However, the present results show the disappearance of this room temperature maximum at higher
strains, and it is thought that this could be due to the
increased influence of the profuse deformation twinning
on work hardening at temperatures below room temperature. At large strains the influence of twinning on
work hardening is thought to be due to the static
hardening effect of twin boundaries acting as deformation barriers [8,20].
Fig. 6 illustrates the engineering stress–strain curves
for the Fe–Ni–C alloy as a function of temperature.
The curves are separated into two groups by different
deformation mechanisms and this is also reflected in the
work hardening behaviour presented in Fig. 7. At small
plastic strains B0.08 the low temperature hardening is
high due to stress-assisted martensite formation which
at − 50°C, near the Ms, has caused large serrations
before yield on the stress-strain curve. At lower test
V. Tsakiris, D.V. Edmonds / Materials Science and Engineering A273–275 (1999) 430–436
433
Fig. 5. Dark-field electron micrographs of banded structure in high-Mn austenite using: (a) 111M, and (b) 111T reflections; (c) diffraction pattern
and (d) analysis (triangular symbols indicate the position of hcp o-martensite reflections if present).
Fig. 6. Engineering stress–strain curves for high-Ni austenite tested at
various temperatures.
Fig. 7. Temperature dependence of work hardening at different true
plastic strains for high-Ni austenite.
434
V. Tsakiris, D.V. Edmonds / Materials Science and Engineering A273–275 (1999) 430–436
temperatures, B Ms, the reduction in available austenite is thought to minimise serrations [21]. This stress-assisted broad lenticular plate-like bcc martensite is
illustrated by Fig. 8. Static hardening of the austenite
by the martensite plates coupled with the hardness of
the bcc martensite itself dominates the mechanical behaviour and tensile ductility is limited. At room temperature (near the upper temperature limit for
stress-assisted martensite, M ss [22]), and above, (with
Md around 100°C) the deformation behaviour is
thought to be dominated by the austenite. The fine
serrations in the stress – strain curve after yielding apparent at 0 and 100°C are consistent with (111) deformation twinning (Fig. 9) but evidence for significant
strain-induced martensite below 100°C was also found,
although saturation magnetisation measurements indicated B 20% (even lower amounts have been measured
by others [12,13]) allowing austenite slip and twinning
mechanisms to dominate. Identification of the strain
bands as deformation twinning confirms previous work
[14,23] but differs from others [12,13,15] who ascribed it
to strain-induced martensite, however, these studies
were either carried out close to M ss or misinterpreted
the diffraction evidence [23]. Fig. 9 is from a specimen
deformed at 100°C where no alternative evidence for
martensite formation was observed. It is also noticed
that the total elongation exhibits a maximum at 100°C
and this may be attributed to enhancement of uniform
elongation by the increased work hardening due to the
profuse deformation twinning.
A comparison of the room temperature deformation
in the high-Mn and high-Ni alloys shows them both to
exhibit serrated flow and to have equivalent work hardening up to a plastic strain of 0.06. This is consistent
with deformation twinning in the austenites, confirmed
to occur, although there is the possibility of strong
dynamic strain ageing in one alloy [10] and strain-induced martensite in the other.
Fig. 8. Deformation microstructure in high-Ni austenite strained to fracture at: (a) − 40°C, light micrograph, and (b) − 20°C, electron
micrograph.
Fig. 9. Banded structure in high-Ni austenite strained to fracture at 100°C: (a) light micrograph, and (b) electron micrograph.
V. Tsakiris, D.V. Edmonds / Materials Science and Engineering A273–275 (1999) 430–436
435
The simulated TRIP steel has a low Ms ( −196°C)
but relatively high Md (35°C). The UTS shows a strong
temperature dependence beneath room temperature
(Fig. 10) characteristic of metastable austenite [24]
which is a reflection of the high work hardening (Fig.
11). Magnetic measurements indicated strain-induced
martensite and evidence for this was also found metallographically as shown in Fig. 12, which is similar to
the appearance found by others [17]. Electron diffraction studies confirmed bcc martensite. The mechanical
behaviour is also not dissimilar to that previously
recorded and explained through the influence of straininduced martensite alone [17,25]. However, in the
present study fine bands similar in morphology to those
found in the other alloys were also detected as shown in
Fig. 13 and identified as (111) deformation twins.
4. Summary
Fig. 10. UTS and yield strength as a function of temperature for
complex-alloyed austenite (TRIP steel).
Fig. 11. Temperature dependence of work hardening at different true
plastic strains for complex-alloyed austenite.
Mechanical behaviour in a range of highly-alloyed
austenites is shown to be influenced by deformation
twinning as well as deformation-induced martensite
transformation. Deformation twinning is operative in a
high-Mn Hadfield steel over a broad temperature and
strain range, and can combine with any unique strain
ageing effects to result in the characteristic high work
hardening. In a high-Ni austenite with Ms and Md
temperatures spanned by the test temperature range an
influence of both stress-assisted and strain-induced
martensite, along with deformation twinning, is found.
In the austenite of a complex-alloyed TRIP steel with
Md just above room temperature the mechanical behaviour at room temperature and below is strongly
influenced by strain-induced martensite although deformation twinning was still evident.
Fig. 12. Deformation microstructure in complex-alloyed austenite strained to fracture at −25°C: (a) light micrograph and (b) electron
micrograph.
436
V. Tsakiris, D.V. Edmonds / Materials Science and Engineering A273–275 (1999) 430–436
Fig. 13. Banded structure in complex-alloyed austenite strained to fracture at room temperature: (a) light micrograph, (b) electron micrograph,
(c) diffraction pattern and (d) analysis.
References
[1] L.E. Murr, K.P. Staudhammer, S.S. Hecker, Metall. Trans. 13A
(1982) 627.
[2] K.P. Staudhammer, L.E. Murr, S.S. Hecker, Acta Metall. 31
(1983) 267.
[3] P. Maulik, J. Burke, A.W. Thompson, Scr. Metall. 17 (1983)
233.
[4] H.M. Otte, Acta Metall. 5 (1957) 614.
[5] C.H. White, R.W.K. Honeycombe, J. Iron Steel Inst. 200 (1962)
457.
[6] W.N. Roberts, Trans. AIME 230 (1964) 372.
[7] Z. Nishiyama, M. Oka, H. Nakagawa, Trans. JIM 6 (1965) 88.
[8] K.S. Raghavan, A.S. Sastri, M.J. Markinkowski, Trans. AIME
245 (1969) 1569.
[9] H.J. Kestenbach, Metallography 10 (1977) 189.
[10] Y.N. Dastur, W.C. Leslie, Metall. Trans. 12A (1981) 749.
[11] T. Maki, S. Shimooka, M. Umemoto, I. Tamura, Trans. JIM 13
(1972) 400.
[12] P.C. Maxwell, A. Goldberg, J.C. Shyne, Metall. Trans. 5 (1974)
1305.
[13] P.C. Maxwell, A. Goldberg, J.C. Shyne, Metall. Trans. 5 (1974)
1319.
[14] H. Onodera, I. Tamura, Scr. Metall. 11 (1977) 1057.
[15] T.N. Durlu, Scr. Metall. 15 (1981) 689.
[16] V.F. Zackay, E.R. Parker, D. Fahr, R. Busch, Trans. ASM. 60
(1967) 252.
[17] G.B. Olson, M. Azrin, Metall. Trans. 9A (1978) 713.
[18] V. Tsakiris, PhD Thesis, University of Oxford, 1986.
[19] L. Remy, Acta Metall. 26 (1978) 443.
[20] L.E. Murr, F.I. Grace, Trans. AIME 245 (1969) 2225.
[21] I. Tamura, T. Maki, H. Hato, Trans. Jap. ISI 10 (1970) 163.
[22] G.F. Bolling, R.H. Richman, Scr. Metall. 4 (1970) 539.
[23] A.K. Sachdev, M.M. Shea, Metall. Trans. 16A (1985) 445.
[24] J.P. Bressanelli, A. Moskowitz, Trans. ASM. 59 (1966) 223.
[25] G.R. Chanani, V.F. Zackay, E.R. Parker, Metall. Trans. 2
(1972) 133.